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Article
A brief review on frictional pressure drop reduction studies for laminar and turbulent flow in helically coiled tubes
Fsadni, Andrew, Whitty, Justin and Stables, Matthew
Available at http://clok.uclan.ac.uk/19602/
Fsadni, Andrew ORCID: 0000-0003-3047-2714, Whitty, Justin ORCID: 0000-0003-1002-5271 and Stables, Matthew ORCID: 0000-0002-9971-9458 (2016) A brief review on frictional pressure drop reduction studies for laminar and turbulent flow in helically coiled tubes. Applied Thermal Engineering, 109 (Part A). pp. 334-343. ISSN 1359-4311
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Accepted Manuscript
A brief review on frictional pressure drop reduction studies for laminar and
turbulent flow in helically coiled tubes
Andrew Michael Fsadni, Justin P.M. Whitty, Matthew A. Stables
PII: S1359-4311(16)31422-3
DOI: http://dx.doi.org/10.1016/j.applthermaleng.2016.08.068
Reference: ATE 8867
To appear in: Applied Thermal Engineering
Received Date: 10 June 2016
Revised Date: 10 August 2016
Accepted Date: 11 August 2016
Please cite this article as: A.M. Fsadni, J.P.M. Whitty, M.A. Stables, A brief review on frictional pressure drop
reduction studies for laminar and turbulent flow in helically coiled tubes, Applied Thermal Engineering (2016), doi:
http://dx.doi.org/10.1016/j.applthermaleng.2016.08.068
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Title: A brief review on frictional pressure drop reduction studies for laminar 3
and turbulent flow in helically coiled tubes 4
5
6
7
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Authors: Andrew Michael Fsadni*, Justin P.M. Whitty, Matthew A. Stables 9
10
*Corresponding author 11
12
Contact details: 13
14
Address: University of Central Lancashire, School of Engineering, Rm. KM124, Preston, 15
UK, PR1 2HE 16
17
Email: [email protected] 18
19
Tel: +44 1772893812 20
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A brief review on frictional pressure drop reduction studies for laminar and turbulent 23
flow in helically coiled tubes 24
25
Abstract 26
27
This review, summarises the pertinent literature on drag reduction (DR) in laminar and 28
turbulent flow in coiled tubes. Due to their compact design, ease of manufacture and superior 29
fluid mixing properties, helically coiled tubes are widely used in numerous industries. 30
However, flow through coiled tubes yields enhanced frictional pressure drops and thus, drag 31
reduction is desirable as it can: decrease the system energy consumption, increase the flow 32
rate and reduce the pipe and pump size. The main findings and correlations for the friction 33
factor are summarised for drag reduction with the: injection of air bubbles and addition of 34
surfactant and polymer additives. The purpose of this study is to provide researchers in 35
academia and industry with a concise and practical summary of the relevant correlations and 36
supporting theory for the calculation of the frictional pressure drop with drag reducing 37
additives in coiled tubes. A significant scope for future research has also been identified in 38
the fields of: air bubble and polymer drag reduction techniques. 39
40
Keywords: Helically coiled tube, drag reduction, frictional pressure drop, surfactants, 41
polymer solutions. 42
43
1. Introduction 44
45
Due to their compact design, ease of manufacture and high efficiency in heat and 46
mass transfer, helically coiled tubes are widely used in a number of industries and processes 47
such as in the food, nuclear, aerospace and power generation industries and in heat recovery, 48
refrigeration, space heating and air-conditioning processes. Due to the formation of a 49
secondary flow, which inherently enhances the mixing of the fluid, helically coiled tube heat 50
exchangers are known to yield improved heat transfer characteristics when compared to 51
straight tube heat exchangers. The secondary flow, which finds its origins in the centrifugal 52
force, is perpendicular to the axial fluid direction and reduces the thickness of the thermal 53
boundary layer. However, for single and multiphase flows, the secondary flow yields a 54
substantial increase in the frictional pressure drop, which often results in diminished system 55
efficiencies (due to enhanced pumping power requirements). For air-water two-phase bubbly 56
flow in helically coiled tubes, Akagawa et al. (1971) reported frictional pressure drops in the 57
range of 58
59
60
3
Figure 1: Schematic representation of helical pipe characteristics. 61
1.1 to 1.5 times greater than those in straight tubes, ceteris paribus, whilst, with the use of 62
nanofluids, such a penalty could nullify the enhanced efficiencies gained with the dispersion 63
of nanoparticles in the base fluid (Aly, 2014). Moreover, due to the secondary flow, the flow 64
characteristics are significantly different to those in straight tubes. Whereas in straight tubes 65
the transition from laminar to turbulent flow occurs at Reynolds numbers in the region of 66
2500, the transition in curved tubes takes place at higher Reynolds numbers. The critical 67
Reynolds number (Eq. (1)) is used to determine the transition of the flow from laminar to 68
turbulent flow (Ito, 1959). 69
70 ������ = 24��.�� (1) 71
72
where δ is the curvature ratio defined through Eq. (2). 73
74
� = ���� (2) 75
76
For δ-1 <8.6E2 whilst for δ-1 >8.6E2, Recrit for a curved tube is equal to that for a straight 77
pipe. 78
79
Another dimensionless number, unique to coiled tubes, is the Dean number, given in 80
Eq. (3). It is used to characterise the flow in curved tubes and quantifies the magnitude of the 81
secondary flow due to the centrifugal force (Mohammed and Narrein, 2012). 82
83
�� = ��√� (3) 84
85
The performance of coiled tubes is a complex function of the coil design parameters 86
(Fig. 1) as well as the resultant pressure drop. Therefore, drag reduction (DR) techniques 87
could be particularly beneficial for systems with curved tubes. Intriguingly, whilst numerous 88
investigations have been reported on DR in straight channels and pipelines with the: injection 89
of air bubbles (Nouri et al., 2013; Fujiwara et al., 2004), dispersion of surfactants (Gasljevic 90
and Matthys, 1997) and polymers (Wei and Willmarth, 1992; Al-Sarkhi and Hanratty, 2001), 91
there is a paucity of research in the field of curved tubes. Moreover, researchers have 92
reviewed the frictional DR techniques in straight channels and pipes (Merkle and Deutsch, 93
1992; Al-Sarkhi, 2010; Murai, 2014) whilst the sole study that reviewed DR in curved tubes 94
was presented by Broniarz-Press et al. (2007). However, the latter focussed on the application 95
of DR surfactant and polymer additives and hence, did not provide a holistic review of the 96
relevant studies. The aim of the current study is to critically review the experimental and 97
numerical studies done on DR in single-phase (water) laminar and turbulent flow through 98
coiled tubes. Such studies are categorized in three sections, representing the pertinent 99
techniques reported. Moreover, this paper complements the earlier review undertaken by the 100
authors of the present study (Fsadni and Whitty, 2016), as it further elucidates the 101
underpinning physics of air-water bubbly flow through curved tubes. It is the authors’ hope 102
that this review will be useful to both academics and industry based engineers through the 103
provision of a concise report on the relevant current knowledge. 104
105
2. Injection of air bubbles 106
107
Over the past 40 years, the injection of microbubbles in the turbulent boundary layer 108
has been investigated by numerous investigators, with the first study reported by McCormick 109
4
and Bhattacharyya (1973) who investigated the DR to a submersible hull. As summarised in 110
Table 1, Shatat et al. (2009a&b) were the first to investigate DR with the injection of air 111
bubbles in laminar and turbulent low through helically coiled tubes. They reported a 112
diminished DR efficiency (Eq. (4)) over that of straight tubes. Such results were more 113
significant with higher curvature ratios whilst, the DR increased with higher air volumetric 114
void fractions (VF) and decreased with higher Re numbers (Fig. 2). Moreover, DR was 115
limited to turbulent flow. Similar results were reported by Saffari et al. (2013) who measured 116
a 25% DR at a VF of 0.09 in turbulent flow bubbly flow. The latter study did not investigate 117
the DR with straight tubes. However, their experimental parameters are comparable to those 118
used by Nouri et al. (2013) who reported a DR of 35% for a VF of 0.09 in straight tubes. 119
�� = 100��������� � (4) 120
121
where fl is the Fanning friction factor for single-phase flow and ftp is the friction factor for 122
two-phase flow. 123
124
For a straight vertical pipe, Fujiwara et al. (2004) reported that, with a high VF in the 125
near-wall region, the turbulence intensity and Reynolds stress are reduced in a wide region of 126
the pipe. The turbulence energy dissipation occurs around the bubbles due to bubble-induced 127
eddies, whilst the diminished fluid density in the near-wall region reduces the shear stress, 128
thus resulting in a lower system frictional pressure drop. Saffari et al. (2013) reported that in 129
curved tubes, higher Re numbers and curvature ratios, result in larger centrifugal forces 130
which force the lower density phase (air bubbles) to migrate towards the inner tube wall 131
region. Resultantly, the shear stress at the inner tube wall region is lower than that at the outer 132
wall region. Hence, the uneven distribution of the air bubbles at higher Re numbers and 133
curvature ratios results in a diminished DR efficiency. 134
135
136
Figure 2: DR as a function of the air VF (α) for a curvature ratio of 0.025 (Shatat et al., 2009a. Fig. 11). 137
These studies are in a general agreement with relevant theory and numerous DR 138
studies reported for channel and straight tube flow. Moreover, there is significant scope for 139
further research in DR (in coiled tubes) as a function of the bubble diameter. In fact, for 140
5
straight tubes and channels, some controversy surrounds the impact of bubble size on the DR, 141
where some investigators reported the DR to be a strong function of the bubble diameter (Liu 142
1993; Murai et al., 2007) while other investigators reported the DR to be independent of the 143
bubble diameter (Moriguchi and Kato, 2002; Shen et al., 2006). The relation of the bubble 144
induced DR studies with those reviewed for two-phase gas-liquid frictional pressure drop 145
characteristics in coiled tubes (Fsadni and Whitty, 2016) remains indeterminate. In fact, the 146
latter investigations reported a general agreement with the Lockhart and Martinelli 147
correlation for straight tubes, with the two-phase frictional pressure drop multiplier in excess 148
of unity. 149
150
3. Surfactant additives 151
152
Surface-active agents (surfactants) are low molecular weight, viscous, non-polymer, 153
water-based chemicals that tend to accumulate at a surface and diminish interactive forces 154
between the molecules of the base fluid, thus reducing the surface tension. Inaba et al. (2005) 155
reported that surfactant additives form a network structure of rod-like micelles which absorbs 156
the turbulent energy with its flexibility and deformation, thus leading to a flow laminarisation 157
effect. Hence, surfactants enhance the elastic properties of the fluid with the resultant 158
increase in DR. Unlike polymer based fluids, the mechanical degradation of the micelle 159
network at high shear stresses is completely reversed at a low flow rate. All the studies 160
reviewed reported a DR limited to the transition and turbulent flows, with a reduced DR in 161
curved tubes when compared to straight tubes, ceteris paribus. Such findings were attributed 162
to the formation of the secondary flow which is largely unaffected by the surfactant additive. 163
Gasljevic and Matthys (1999) reported that for a velocity range of 2-5m/s, the secondary flow 164
effects were separated from the turbulence effects through the use of the turbulence reduction 165
– drag (TRD) method given in Eq. (5). This yielded a TDR of 70% (turbulence suppression) 166
for both coiled and straight tubes (Fig. 3). In contrast, Broniarz-Press et al. (2003) reported 167
that the tube curvature effect on the friction factor was diminished due to the damping of the 168
secondary flows streams. A broad analogy can be made with nanofluid flow in coiled tubes 169
where, nanoparticles were also attributed to the mitigation of the secondary flow (Fsadni and 170
Whitty, 2016). 171
172
��� = � !",�!�� $%&� !",�!�� !",�' (5) 173
174
where lm refers to the laminar flow of the base fluid (without the DR additives) at the same 175
Re number and tb refers to the turbulent flow of the base fluid. 176
6
177
Figure 3: Friction reduction in terms of DR and TRD for a coiled and straight pipe (Gasljevic and 178
Matthys, 1999 Fig. 4). 179
At laminar flow conditions, Weber et al. (1991) and Gasljevic and Matthys (2009) 180
reported an increase in the frictional pressure drop (compared to water). This was attributed 181
to the enhanced solution viscosity. There is a general agreement amongst the studies 182
reviewed that lower coil curvatures and higher surfactant concentrations yielded higher DR 183
efficiencies. Moreover, Kamel and Shah (2013) reported that at higher concentrations, 184
surfactant solutions are more resistant to mechanical degradation and hence, yield higher DR 185
efficiencies at increased Re numbers. Therefore, Broniarz-Press et al. (2002) reported that 186
DR is a strong function of the surfactant concentration, with DR evident above a critical 187
concentration. Inaba et al. (2005) reported that the dynamic nature of surfactant DR additives 188
render them particularly relevant for heating systems. However, such comments should be 189
considered in light of the fact that these additives are known to yield reduced heat transfer 190
coefficients. Kostic (1994) attributed this phenomenon to the non-homogenous turbulence 191
resulting from the flow-induced anisotropicity of the highly structured micelle network. 192
Weber et al. (1991), Inaba et al. (2000&2005), Aly et al. (2006) and Kamel and Shah (2013) 193
presented correlations for the calculation of the friction factor in surfactant solutions. Due to 194
the Non-Newtonian properties of these solutions (C>3,000ppm), correlations were developed 195
as a function of the modified or generalised Re and De numbers. 196
197
4. Polymers additives 198
199
Toms (1948) reported that the addition of minute concentrations of high-molecular 200
weight, long chain and flexible polymers to a Newtonian solvent can yield significant DR 201
properties. Whilst it is widely accepted that the DR efficiency is a strong function molecular 202
weight and distribution, molecular structure and solubility, the underpinning physics are 203
known to be complex and not well-understood (Gallego and Shah, 2009). Factors such as 204
shear thinning, viscoelasticity and molecular stretching have been suggested to diminish the 205
turbulence in the fluid (Bird et al., 1987), thus resulting in DR. 206
Shah and Zhou (2001) stated that the DR mechanism of polymers occurs at the 207
boundary layer and therefore is typically more effective in smaller tube diameters. Moreover, 208
7
in agreement with the findings reported for air-bubble injection, DR efficiency decreases with 209
higher coil curvatures. This is inherent to the effects of the centrifugal force on the fluid 210
flow. DR is also a function of the ability of the polymer to resist thermal and mechanical 211
degradation. Shah et al. (2006) reported that at a volume concentration of 0.07%, the widely 212
used partially hydrolysed polyacrylamide (PHPA) copolymer (Nalco ASP-820) yielded the 213
highest DR (65%). At this concentration, it was assumed that the fluid behaviour is quasi-214
Newtonian. This concentration was subsequently used by Gallego and Shah (2009) and 215
Ahmed Kamel (2011). Gallego and Shah presented a unique generalised friction pressure 216
correlation for DR polymer solutions in coiled tubes. Their correlation assumed that the 217
appropriate characteristic polymer solution viscosity is relative to the zero shear rate 218
viscosity, that is, the shear stress required to deform the polymer molecule from its 219
equilibrium state. 220
The effect of the polymer concentration is also function of the specific physical 221
conditions of the flow. Resultantly, Shah and Zhou (2001) reported that for large tubes and 222
low flow rates, high concentrations of polymer additives increased the fluid drag and delayed 223
the onset of DR (Fig. 4). For small diameter tubes, the opposite effect was reported and thus, 224
a higher polymer concentration increased the DR. 225
226
227 Figure 4: Effect of polymer concentration (Xanthan) on DR ratio (Shah and Zhou, 2001 Fig. 5). 228
The effect of elevated temperatures on the DR of polymers in coiled tubes was 229
investigated by Gallego and Shah (2009) and Ahmed Kamel (2011) who reported that, in 230
contrast to the findings for straight tubes, DR remained quasi-constant (Ahmed Kamel) or 231
increased (Gallego and Shah) with temperature. It is widely accepted that with polymer 232
solutions in straight tubes, elevated temperatures yield a drop in the DR. This is due to a 233
combination of factors, such as the deterioration of the solvent-polymer interaction and the 234
diminishing of the macromolecule size (Clifford and Sorbie, 1985; Nesyn et al., 1989). In 235
view of this complexity and the paucity of studies for curved tubes, Gallego and Shah (2009) 236
and Ahmed Kamel (2011) concluded that the origins of their results are indeterminate and 237
thus require further investigation. In contrast to the numerous studies on polymer DR 238
additives to gas-liquid flows in straight tubes (Sylvester and Brill, 1976; Al-Sarkhi and 239
8
Soleimani, 2004), there are no related studies for coiled tubes. This presents further scope for 240
future research in the field of two-phase flow in coiled tubes. 241
242
Investigators
&
Methodology
Year Flow configuration &
coil geometry
Mean bubble
size
Void fraction
or
concentration
Drag reduction
Air bubbles
Shatat et al.
Experimental
2009a
&b
dt=20mm Dc=800,400,200mm
δ=0.025,0.05,0.1 H=40mm
1,000<Re<100,000 We<1.0
Laminar and turbulent
bubbly flow
db,m=0.06mm
db,max=0.174m
m
No
deformation of
bubbles.
0.21<VF<0.44%
16% for δ=0.025. For a
straight pipe 51% DR,
ceteris paribus. DR effect starts at the
critical Re number.
DR increases with VF
for all cases. The curvature of the coils had a negative
effect on drag reduction.
The Re number corresponding to the
maximum DR was
shifted to a higher value (compared to a straight
tube). This shift increased with an
increase in the curvature of the coil.
Saffari et al.
Experimental
2013 dt=12,19mm
Dc=200mm δ=0.06,0.095
H=24mm
P=0.101MPa 10,000<Re<50,000
Turbulent bubbly flow
db,m=0.27mm
Bubble
diameter
decreased at
higher Re
numbers. At
lower Re
numbers,
bubbles were
less spherical
in shape (less rigid). This is
due to the
influence of
flow stress and
reduced
surface
tension (in
comparison to
the smaller
bubbles).
0.01<VF<0.09
DR increased with
VF with a maximum
of 25% at a VF of
9%. DR diminished
with higher Re
numbers.
At a low VF of 1%, a
DR of 9% was
measured.
DR diminished with
an increase in the curvature of the coil.
Saffari and
Moosavi
Numerical
(Eulerian-
Eulerian
multiphase
model)
2014 dt=16,25,40mm Dc=100,200mm
δ=0.08,0.125,0.20 H=20,60
15,000<Re<80,000
Turbulent bubbly flow
db,m=0.1mm
No
deformation of bubbles.
0.01<VF<0.09
Due to a reduction in
the mixture density,
higher VF yields lower pressure drops,
shear stress and
friction coefficient.
9
Surfactant solutions & Foam fluids
Weber et al.
Experimental
1991 dt=10.5,16.5mm 157<Dc<454mm
0.105<δ<0.036, N=12,18,34,39
1,500<Re<100,000
6,750<Recrit<9,480
30oC<T<90oC
Laminar and turbulent
Fluid was
assumed to be
quasi-
Newtonian.
C=62.5;250;1,
000 ppm
Habon in
water.
For laminar flow,
surfactant additives
increased the fluid
drag. For turbulent flow the
increase in DR with
C was marginal.
DR in curved tubes
diminished at a lower
Re value than that in
straight tube, ceteris
paribus.
(�)**�*+ = 1855����� + 0.011
Gasljevic and
Matthys
Experimental
1999 dt=2mm Dc=200mm
δ=0.01 1.8<V<7m/s
T=25oC
Laminar and turbulent
Fluid was
assumed to be
quasi-
Newtonian.
C=2,000ppm
SPE95285
(Same
viscosity as
water)
DR in coiled tube is
30%, in a straight
tube 60%, ceteris
paribus.
Calculated 70%
reduction in turbulence effects for
both straight and
coiled tubes.
At V>5m/s DR effect
diminishes due to
micelle degradation.
Inaba et al.
Experimental
2000 dt=17.7mm
Dc=177,300.9,442.5,885mm
δ=0.02,0.04,0.059,0.1 400<Re’<200,000
10oC<T<25oC
θ=45o,90o,180o,270o
Laminar and turbulent
Non-
Newtonian
viscoelastic
fluid.
530<C<1,773
ppm
Dodecyltrimet
hyl
Ammonium Chloride
(C12H25N(CH3
)3 =263.89)
and Sodium
Salicylate
(C7H5NaO3=1
60.10) in
water
No DR at laminar
flow conditions,
whilst DR at
turbulent flow
conditions was less in relation to that in a
straight pipe.
At a C of 561ppm no
DR was measured.
Due to the
suppression of
turbulence vortexes,
the heat transfer
coefficient was less
than that for water.
(�)��/ = 6.75 2��3� 4��.56� 7�.896��′��.5
0.02<δ<0.05; 45o<θ<270o; C>1,000ppm
(SD=9.17%)
Broniarz-Press
et al.
Experimental
2002 0.0219<δ<0.0792 1,200<Regen<30,000
70<De’’<3,000 T=303,323,333K
Laminar and turbulent
Non-
Newtonian
viscoelastic
fluid.
WC=0.1,0.25
%
Cationic
Hexadecyltrim
ethylammoniu
m chloride
(HTAC) and
DR is only evident
above a critical C.
This contrasts to
polymers where DR
is significant with
minute C of polymer
additives.
10
anionic soaps,
sodium &
potassium
oleates with
WC=2.5,7%
sodium
salicylate
(NaSal),
sodium
chloride, and
potassium
chloride
solution
additives in
water.
With polymer
additives, DR is only
evident when the
molar mass is above a
critical value.
Cylindrical micelles
stabilise the
mechanisms of
curved flow.
DR increases with
higher turbulence.
Broniarz-Press
et al.
Experimental
2003 0.0219<δ<0.0792 1,200<Regen<30,000
70<De’’<3,000 T=303,313,333K
Laminar and turbulent
Non-
Newtonian
viscoelastic
fluid.
WC=0.1,0.25
%
Cationic
Hexadecyltrim
ethylammonium chloride
(HTAC) and
anionic soaps,
sodium &
potassium
oleates with
WC=2.5,7%
sodium
salicylate
(NaSal),
sodium chloride, and
potassium
chloride
solution
additives in
water.
DR observed in
turbulent and
pseudolaminar flows.
Surfactant additives
diminished the tube curvature effect on
the friction factor.
This was attributed to
the damping of the
secondary flow
streams.
Inaba et al.
Experimental
2005 dt=14.4mm
Dc=540mm δ=0.0267
H=32mm
N=10 10,000<Re’<100,000
100<De/De’<10,000 100<Gz/Gz’<10,000
5oC<T<20oC Laminar and turbulent
Non-
Newtonian
viscoelastic
behaviour at
high
concentrations (>3,000ppm)
1,000<C<3,50
00ppm
Mixture of
oleyldihydrox
yethylamineox
ide (ODEAO, C22H45NO3=3
71) 90%, non-
ionic
surfactant &
cetyldimethyla
minoaciticacid
betaine
(CDMB,
C20H41NO2=3
27) 10% as a
zwitterion
surfactant in water.
43% DR in the coiled
tube.
77% DR in a straight
tube.
This is due to the
secondary flow that contributes towards
the pressure drop in
coiled tubes.
Drop in the heat
transfer coefficient
with surfactant C.
DR increases with
surfactant C.
11
(�,�)��/(;�,�)��/ = ��<�.9�=*��.88�*�8.5
where:
�*� = >?��@?�>�AB�B�?�(DEFG); =*� = ?��@?�
�AB�B�?�(J,KKK��')
Aly et al.
Experimental
2006 dt=14.4mm Dc=320,540,800,mm
0.018<δ<0.045 H=32mm
N=10
1,000<Re’<100,000 5oC<T<20oC
Laminar and turbulent
Newtonian
fluids for
C<3,000ppm.
250<C<5,000
ppm
Mixture of
non-ionic
surfactant oleyldihydrox
yethylamineox
ide (ODEAO,
C22H45NO3=3
71) 90%, &
cetyldimethyla
minoaciticacid
betaine
(CDMB,
C20H41NO2=3
27) 10% as a
zwitterion surfactant in
water.
DR increased with
surfactant C, with a
max. of 59% at
Re’=55,350 and
C=2678ppm. DR increased with
temperature and
decreased with higher
coil curvatures.
Lower DR and losses
in the heat transfer
coefficient were
measured when
compared to straight
tubes, ceteris paribus.
(�)��/ = 137��.6�(1 + 0.94=N��.�9�N�8.5O)(1.56 + PQR��′)5.O�
(SD=10%)
1<Tc<1.065; 4<Cc<14; 0.018<δ<0.045
Gasljevic and
Matthys
Experimental
2009 dt=12mm
δ=0.043,0.067,0.116 0.9<V<7m/s
T=25oC
Laminar and turbulent
Non-
Newtonian
viscoelastic
fluid.
C=2,000ppm
cationic
surfactant
Ethoquad T-
13 &
2,000ppm
NaSl as a counterion.
DR for turbulent flow
in the range of 30-
40% was measured.
This is less that that
in a straight pipe
where 75% DR was
measured, ceteris paribus.
DR decreased with
higher curvature
ratios.
For the coil with the
highest curvature, at
V=0.9m/s, the
pressure drop
increased in relation
to that of water. This
was attributed to the
higher viscosity of the surfactant
solution in relation to
water at a shear rate
of 500s-1
.
Kamel and
Shah
Experimental
2013 11.0<dt<63.5mm 360<Dc<2,850mm
0.01<δ<0.031 20,000<Re<200,000
Turbulent
Non-
Newtonian
viscoelastic
fluid.
VC=1.5,2.3,4
%
Tallowalkyla
midopropyl
DR is significant in
coiled tubes and
increases with C,
with a significant
12
dimethylamine
oxide
viscoelastic
surfactant
(VES)
containing 50-
65% WC
active
surfactant, 25-
40%
propylene
glycol and
water as
solvents.
increase above a VC
of 2%. Higher C also
exhibit higher
resistance to
mechanical
degradation.
Surfactant based
fluids are more
resistant to shear
degradation than
polymer based fluids.
Larger tube diameters
and smaller curvature
ratios yield larger
DR.
(�)**�*+ = (−32,200.42�� + 1,830.62�� + 0.32)��+T*UO,�8�.V5WX��86.VOW��.55Y
where:
��+T* = Z3�*[��*\8*�8] ^
Wang et al.
Numerical
2015 dt=7.3mm
Dc=203mm δ=0.036
V=3m/s
Compressible
Non-
Newtonian
foam fluid.
65<Γ<98 The secondary flow
effect (vortex roll) of
the foam fluid is
smaller than that of
water.
Polymer solutions
Barnes and
Walters
Experimental
1969
dt=8,9.6mm 60<Dc<3000mm
0<Q<80cm3/s T=20oC
Spiral coil Laminar and turbulent
Non-
Newtonian
viscoelastic
fluid.
Solvent: Water
VC=0.025,0.0
3,0.05,0.10%
Polyacrylamid
e (P250);
Polyethylene oxide (Polyox
SR305) and
Guar Gum.
Easier to pump
viscoelastic liquids in
curved tubes.
Suppression of
turbulence with polymer additives
which renders the
flow almost laminar.
Curvature enhances
DR in the transition
region, whilst it
reduces DR at high
Re numbers.
Kelkar and
Mashelkar
Experimental
1972 dt=12.5mm
Dc=665mm δ=0.019
H=38mm N=6
10<Re<100,000
Laminar and turbulent
Non-
Newtonian
viscoelastic
fluid. Solvent:
Water
50<C<500pp
m
Polyacrylamid
e (AP30&ET59
7)
0.76<n<1.00
DR limited to
turbulent flow. DR
increases with
polymer C up to a critical Re when DR
diminishes.
_ = 0.2 + 0.81 + (`�T< )�.a
where:
�̀T< = � b$��cTK.EF
Z� b$��cTK.EF^dAeK.f
; _ = �.6 ;�
Mashelkar and
Devarajan
Experimental
1976 dt=12.48,12.49,12.50mm 92.3<Dc<1,282mm
0.01<δ<0.135 H=38.1mm
3<N<40
Non-
Newtonian
viscoelastic
fluid. Solvent:
0.01<C<0.5%
Carboxymethy
l cellulose
(CMC), Polyacrylamid
The PEO and PAA
polymer yielded the
best DR, even at the
lowest C. This was attributed to the fluid
13
10<Regen<100,000 70<De<400
40<Wi<950 Laminar and turbulent
Water e (PAA-AP-
30)
0.354<n<0.99
Polyethylene
oxide (PEO-
WSR-301)
0.871<n<0.99
elasticity.
(g,�)**�*+ = (;(1 − 0.03923hi�.�9aa) where: (;,�)**�*+ = (9.069 − 9.438j + 4.374j�)��.5��′′(��.O6ak�.8��*)
0.35<n<1
Oliver and
Asghar
Experimental
1976 6.72<dt<14.0mm
0.033<δ<0.082 152<L/dt<410
N=3-4 60<De<2,000
10<Gz<400 Laminar
Non-
Newtonian
viscoelastic
fluid.
Solvent:
Water.
250<C<2,500
ppm
Polyacrylamid
e Separan
AP273 in
water and a
56/44 (WC)
glycerol/water
solution with
500ppm
Separan
AP273.
Some DR due to the
partial suppression of
the secondary flow.
Rao
Experimental
1993
dt=9.35mm 98<Dc<247mm
0.038<δ<0.095 H=19.5mm
8<N<20
10,000<Re<60,000 Turbulent
Non-Newtonian
viscoelastic
fluid.
Solvent:
Water
C=50,100,200ppm
Polyacrylamid
e (Praestol
2273TR)
Higher DR with higher polymer C and
smaller coil
curvatures.
Azouz et al.
Experimental
1998 dt=30mm pH=9,10,11
100<Regen<100,000 Laminar and Turbulent
Non-Newtonian
viscoelastic
fluid.
Solvent:
Water
C=35,40 lb/kgal
Linear Guar
gum &
Hydroxypropy
l Guar (HPG),
Crosslinked
Guar gum &
Hydroxypropy
l Guar (HPG)
with 12% sol.
of boric acid
as crosslinking agent.
For borate-crosslinked HPG, the
pressure gradient is a
strong function of pH
and the tube length.
For borate
crosslinked guar, the
pressure gradient is
pH dependent but is
not effected by the
tube length.
14
Shah and
Zhou
Experimental
2001 dt=25.4,38.1,60.3mm Dc=121.92,182.88,281.94
mm δ=0.0113,0.0165,0.0169
Pmax=34.47MPa 4,000<Regen<200,000
Laminar and Turbulent
Non-
Newtonian
viscoelastic
fluid.
Solvent:
Water
Guar
C=2.397
kg/m3
0.642<n<0.72
C=3.595
kg/m3
0.527<n<0.55
C=4.793
kg/m3
0.433<n<0.48
3
partially
hydrolysed
polyacrylamid
e (PHPA),
C= 2.397
kg/m3
0.355<n<0.38
4 C=4.793
kg/m3
0.305<n<0.32
2
Xathan gum
C=1.198
0.472<n<0.48
9
C=2.397
0.381<n<0.43
9 C=4.793
0.277<n<0.34
3
hydroxyethylc
ellulose
(HEC)
C= 2.397
0.6<n<0.668
C=3.595
0.494<n<0.54
5 C=4.793
0.42<n<0.443
DR of polymer
solutions decreases
with the curvature
ratio.
Xathan and PHPA
yielded the best DR
properties. HEC
resulted in no DR.
Higher DR with
smallest tube
diameters.
For the largest tube
diameter, higher
polymer C decreased
the onset of the DR
whilst the opposite
effect was reported
for the smallest tube
diameter.
Shah et al.
Experimental
2006 dt=11mm
Dc=35.60,57.24,109.97mm
δ=0.01,0.019,0.031
N=3,6 22,000<Res<155,000
Turbulent
For
0.01<C<0.07
% fluid is
assumed to be
Newtonian.
Non-
Newtonian
viscoelastic
fluid for
C>0.07%.
Solvent: Water
Nalco ASP-
820 (PHPA)
0.01<VC<0.1
5%
0.814<n<1.00
Optimum VC of
ASP-820 is 0.07%.
At 0.07%, ASP-820
yields a DR of 75%
in straight tube and
65% in coiled tube,
ceteris paribus.
Increase in flow rate
increases the DR
while the opposite
effect was reported for an increase in
curvature.
An increase in the
polymer C or
curvature ratio delays
the onset if DR.
15
(g,�)**�*+ = l<�mn 2 8.�cTopn4 where A’,B’&C’ are constants given in Shah and Ahmed
Kamel, (2005) and is valid for VC=0.07%.
(ME= ±6%)
Zhou et al.
Experimental
2006 dt=11.05mm Dc=12.14,29.67,47.70,91.
64mm δ=0.010,0.019,0.031,0.07
6
N=3,6,7 5,000<Regen<100,000
Laminar and turbulent
Non-
Newtonian
viscoelastic fluid.
Solvent:
Water
C=10,20,30
lb/Mgal
Guar gum, C=10,15,20,30
lb/Mgal
Hydroxypropy
l Guar (HPG),
C=10,20,30
lb/Mgal
Xanthan gum
DR in coiled tubing is
diminished (by 10-
30%) in relation to that in a straight tube,
ceteris paribus.
DR in coiled tubing is
increased with higher
Re. This contrasts to
the case of straight
tubes, where DR
diminishes at higher
Re.
DR increased with C
of Xanthan. Curvature delayed the
onset of DR as a
result of the delay in
the onset of
turbulence.
Gallego and
Shah
Experimental
2009 dt=11,20.57mm
Dc=35.60,57.24,109.97,182.88cm
δ=0.01, 0.0113,
0.019,0.031 22,000<Res<430,000
T=21.1,37.7,54.4oC Turbulent
For
0.01<C<0.07
% fluid is
assumed to be
Newtonian.
Non-
Newtonian viscoelastic
fluid for
C>0.07%.
Solvent:
Water
Nalco ASP-
700 & ASP-
820 (PHPA)
VC=0.05,0.07,
0.10,0.15%
0.75<n<1.00
DR decreases with
curvature.
DR in coiled tubes is
lower than that in
straight tubes, ceteris
paribus. At 0.07%
ASP-820, DR is 77% in a straight tube and
64% in the coiled
tube (79%&59% for
ASP-700).
The increase in T
resulted in a decrease
of DR in straight
tubes. The opposite
effect was measured
in coiled tubes
(DR=45%,52%&55% at 21.1,37.7,54.4
oC
respectively for ASP-
820)
DR decreases with
tube roughness in
both straight and
coiled tubes (64% to
60% for coiled tube).
`�T =qrrrs 1.6675 ∗ 10��u(;,�)**�*+��;v8.9�a9 �8wx3� �Z1 + 1.0974 ∗ 10�� �(;,�)**�*+��; 8wx3� �
8.9���5^�.O588
yzzz{|\g};\g}~�
�.88�V
16
`�T = Z(;,�)**�*+(g,�)**�*+^�− 1
(ME= ±10%)
Shah and
Zhou
Experimental
2009 dt=12mm Dc=146,356,572, 1100
mm δ=0.01,0.019,0.031,0.076
N=3,3,7
3,700<Regen<11,500 Laminar and turbulent
Non-
Newtonian
viscoelastic
fluid.
Solvent:
Water
1.198<C<3.59
5 kg/m3
Guar gum,
0.482<n<0.81
9
Hydroxypropy
l Guar (HPG),
0.485<n<0.80
5
Xanthan gum 0.310<n<0.71
7
Significant DR with
all three polymer
fluids. Curvature
reduces the DR and
delays the onset of
DR.
1�(�)**�*+ =
10.05311 + 0.29465��.5 PQR8� 2��+T*(
8�4 + 10.03094 + 0.24575��.5
Ogugbue and
Shah
Numerical
2011 δ=0.3,0.5,0.6,0.8
ε=0,0.25,0.5,0.75,0.96 100<Regen<10,000
Laminar and turbulent
Non-
Newtonian
viscoelastic
fluid.
Solvent:
Water
C=20,30,40,60
lb/Mgal
Guar
0.335<n<0.66
6
DR increases with
increased eccentricity
(50% reduction for
fully eccentric
annular section)
Higher C increased
the frictional pressure
drop for laminar flow.
For turbulent flow, all
C resulted in a
significant DR.
(�)**�*+ = 0.00378 3T��3�~� +3.7374��+T* + 4042
2��+T* −0.00124
(ME= ±5%)
Ahmed Kamel
Experimental
2011 dt=11mm Dc=579mm δ=0.019
T=22,35,38oC 20,000<Re<200,000
Pmax=6.9MPa Turbulent
Properties
assumed to be
quasi-
Newtonian. Solvent:
Water
Nalco ASP-
820 (PHPA)
VC=0.07%
n ≈ 1.00
DR in the range of
30-80%
At elevated T, the DR
effect is diminished in straight tubes
while it remains
quasi- constant in
coiled tubes.
��>��) = 1.0
(ME= ±2.1%)
Table 1: Review of the experimental and numerical work 243
244
5. Conclusions 245
246
17
The studies reviewed have demonstrated that, due to the secondary flow, which 247
increases with curvature, DR in coiled tubes is diminished when compared to straight tubes. 248
However, a significant DR can be still be achieved with the introduction of: bubbles (9-25%), 249
surfactant (30-59%) and polymer (circa 30-80%) additives. DR is a strong function of the 250
surfactant concentration and the air volume fraction whilst with polymer additives DR 251
efficiency is dependent on the molecular weight, structure and solubility. DR is generally 252
present in flows with Re numbers in excess of the critical number. However, at elevated Re 253
numbers DR diminishes. This is due to the higher centrifugal forces (air bubbles and 254
polymers) and mechanical degradation with high shear stress (surfactants). A number of 255
authors have presented correlations for the calculation of the friction factor which are 256
typically a function of the: curvature ratio, Re and De numbers and the additive 257
concentration. 258
Due to their low molecular weights, viscous properties and resilience to mechanical 259
degradation, surfactant based fluids are generally considered to be superior to polymer based 260
fluids. Hence, surfactants are suitable for a variety of applications such as district cooling and 261
heating systems. A significant scope for future research has been elucidated for DR in coiled 262
tubes with the injection of air bubbles (impact of bubble size and relation with the Lockhart 263
and Martinelli correlation) and the application of a combination of methods, such as the use 264
of polymer and surfactant additives with bubbly flow. 265
266
Acknowledgments 267
268
The authors of the current investigation would like to thank the University of Central 269
Lancashire UK, for facilitating the completion of this study as well as the various authors 270
who have been contacted during the course of this study. 271
272
Notation List 273
274
C concentration (ppm) 275
Cc non-dimensional surfactant concentration (-) 276
Cst empirical constant (-) 277
d tube internal diameter (m) 278
dr drag ratio (-) 279
D helix diameter (m) 280
De Dean number (Reδ1/2
) (-) 281
De’ modified Dean number (Re’δ 1/2
) (-) 282
De’’ modified Dean number (Regenδ1/2
) (-) 283
DR drag reduction (%) 284
f friction factor (-) 285
FC friction coefficient (-) 286
Gz Graetz number (RePr/z) (-) 287
Gz’ modified Graetz number (Re’Pr’/z) (-) 288
H pitch (m) 289
K rheometric and technical consistency index (Pa sn) 290
L length (m) 291
ME mean error (%) 292
n power law model flow behaviour index (-) 293
N number of turns (-) 294
NDe Deborah number (-) 295
NDe’ modified Deborah number (-) 296
18
P pressure (Pa) 297
Pr Prandtl number (-) 298
Pr’ modified Prandtl number (-) 299
Q volume flow rate (m3/s) 300
Re Reynolds number (-) 301
Re’ modified Reynolds number as proposed by Metzner and Reed (1955) 302
�88�* ��*k89* � ��D������� �� (-) 303
Recrit critical Reynolds number (24��.��) (-) 304
Regen generalised Reynolds number ��D������a��J� � (-) 305
SD standard deviation (%) 306
T temperature (0C) 307
Tc non-dimensional surfactant solution temperature (-) 308
TRD turbulence reduction: drag (-) 309
V flow velocity (m/s) 310
VC volume concentration (%) 311
VF volumetric void fraction (-) 312
We Weber number (-) 313
Wi Weissenberg number (σel/σv) (-) 314
WC weight concentration (%) 315
x axial distance of coiled pipe (m) 316
z dimensionless axial distance (x/dt) (-) 317
318
Greek 319
320
β reduced friction factor (-) 321
δ curvature ratio (-) 322
ε coil eccentricity (-) 323
θ angle from inlet of curved pipe (o) 324
λ relaxation time (s) 325
µ viscosity (cP) 326
µo zero shear rate viscosity (cP) 327
ν average fluid velocity (ft/s) 328
ρ density (kg/m3) 329
σ stress (N/m2) 330
Γ quality (%) 331
332
Subscripts 333
334
a ambient temp 335
b bubble 336
bf base fluid 337
c coil 338
crit critical 339
DRF drag reducing fluid 340
eff effective 341
el elastic 342
eit external diameter of inner tubing 343
gen generalised 344
iot internal diameter of outer tubing 345
19
l liquid 346
lm laminar 347
m mean 348
nd non-dimensional 349
o zero 350
p polymer solution 351
s solvent 352
st straight tube 353
t tube 354
tb turbulent 355
tp two-phase 356
T elevated temperature 357
v viscous 358
359
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Highlights
Review on pressure drop reduction studies in helically coiled tubes
Air bubbles, surfactant and polymer additives are effective in diminishing drag
Drag reduction is diminished in relation to straight tubes
Drag reduction is predominantly evident in turbulent flow
Drag reduction diminishes with higher coil curvatures and excessive Re numbers
*Highlights (for review)